Application Report SNVA408B – January 2010 – Revised April 2013 AN-1994 Modeling and Design of Current Mode Control Boost Converters ..................................................................................................................................................... ABSTRACT This application note presents a detail modeling and design of current mode control boost converters operating in the continuous conduction mode (CCM). Based on the derived small signal models, the design of a lag compensator for current mode control boost converters will be detailed. The LM3478 boost controller will be used in the example. Simulation and hardware measurement of frequency responses will be shown. 1 2 3 4 5 6 Contents Basic Operation of a Boost Converter ................................................................................... Modeling of an Open Loop Boost Converter ............................................................................ Modeling of a Current Mode Control Boost Converter ................................................................. Principle of a Lag Compensator .......................................................................................... Illustrative Example ......................................................................................................... Conclusion ................................................................................................................... 2 2 4 6 7 9 List of Figures 1 An Open Loop Boost Converter........................................................................................... 2 2 Inductor Current Waveform at the On Period ........................................................................... 4 3 Frequency Response of a Lag Compensator ........................................................................... 6 4 A Lag Compensator Implemented by a Transconductance Amplifier Circuit ....................................... 6 5 Frequency Response of the Un-Compensated System 6 Frequency Response of the Compensated System with 90° Phase Margin ........................................ 9 ............................................................... 8 List of Tables 1 Major Parameters of the Example Boost Converter .................................................................... 7 2 Parameters of the LM3478 ................................................................................................ 7 All trademarks are the property of their respective owners. SNVA408B – January 2010 – Revised April 2013 Submit Documentation Feedback AN-1994 Modeling and Design of Current Mode Control Boost Converters Copyright © 2010–2013, Texas Instruments Incorporated 1 Basic Operation of a Boost Converter 1 www.ti.com Basic Operation of a Boost Converter Figure 1. An Open Loop Boost Converter Figure 1 shows an open loop boost converter with an inductor L1, a diode D1, an output capacitor COUT with an equivalent series resistance RCOUT. It is assumed that the load is a resistor ROUT, and the switch Q1 is ideal. Let νIN, νOUT, and νCOUT be the input voltage, output voltage, and the voltage across COUT, iL1 be the current through L1, and VD1 be the forward voltage drop of D1 when D1 is turned on. Under the CCM, when Q1 is turned on, the state equations are QIN = L1 QOUT ROUT d i , dt L1 (1) d Q = -COUT dt COUT (2) Also, the output equation is QOUT = QCOUT + COUT d QCOUTRCOUT dt (3) Similarly, when Q1 is turned off, the output equation of (3) still holds, while the state equations become QIN = L1 d i + VD1 + QOUT, dt L1 (4) QOUT d = iL1 - COUT QCOUT dt ROUT 2 (5) Modeling of an Open Loop Boost Converter To obtain a small signal model of boost converters, it is required to apply the averaging technique, perturbation, and the linearization technique. First, by applying the averaging technique, the averaged state equations and output equation are QIN = L1 d i + (1 - d)VD1 + (1 - d)QOUT, dt L1 (6) QOUT d (1 - d)iL1 - COUT QCOUT, dt ROUT = (7) d QOUT = QCOUT + RCOUTCOUT QCOUT dt (8) where d is the duty cycle, x is the averaged variable for the variable x (which can represent νIN, νOUT, νCOUT, and iL1). Second, by applying small signal perturbations to (6) to (8), i.e. let x=X+~ x, ~ where X and x are nominal (DC) and perturbed (AC) variables, d ~ ~ ~ VIN + ~ QIN = L1 (IL1 + iL1) + (1 - D - d)VD1 + (1 - D - d)(VOUT + ~ QOUT), dt 2 AN-1994 Modeling and Design of Current Mode Control Boost Converters (9) SNVA408B – January 2010 – Revised April 2013 Submit Documentation Feedback Copyright © 2010–2013, Texas Instruments Incorporated Modeling of an Open Loop Boost Converter www.ti.com (VOUT + ~ QOUT) ~ ~ d (V +~ Q ), = (1 - D - d)(IL1 + iL1) -COUT dt COUT COUT ROUT VOUT + ~ QOUT = VCOUT + ~ QCOUT + RCOUTCOUT d ~ dt (VCOUT + QCOUT) (10) (11) Third, by applying the linearization technique (assume that the high order non-linear terms are small and negligible), a set of DC and AC equations can be obtained as follows: DC equations: From (9) VIN = (1 - D)VD1 + (1 - D)VOUT D= VOUT - VIN + VD1 . VOUT + VD1 (12) Also VOUT = VIN - (1 - D)VD1 . (1 - D) For simplicity, consider that (1 - D)VD1 is small compared with VIN, VOUT = VIN . (1 - D) (13) From (10), IL1 = VOUT . (1 - D)ROUT (14) AC equations: From (9), ~ ~ ~ ~ vIN = sL1iL1 + (1 - D)Q OUT - dVOUT ~ ~ ~ sL1iL1 = ~ vIN - (1 - D)Q OUT + dVOUT (15) From (10), ~ QOUT ROUT ~ ~ = (1 - D)iL1 - dIL1 - sCOUT~ QCOUT (16) From (11), ~ QOUT = ~ QCOUT + sRCOUTCOUT~ QCOUT, ~ QCOUT = ~Q OUT , 1 + sRCOUTCOUT (17) Substitute (13), (14), (15), and (17) into (16), (1 + sRCOUTCOUT) ~ QIN (1 - D) ~ QOUT = 1+s L1 ROUT(1 - D)2 + (1 + sRCOUTCOUT) VIN (1 - D)2 + RCOUTCOUT + s2 SNVA408B – January 2010 – Revised April 2013 Submit Documentation Feedback 1- sL1 ~ d ROUT(1 - D)2 L1COUT(ROUT + RCOUT) ROUT(1 - D)2 AN-1994 Modeling and Design of Current Mode Control Boost Converters Copyright © 2010–2013, Texas Instruments Incorporated (18) 3 Modeling of a Current Mode Control Boost Converter 3 www.ti.com Modeling of a Current Mode Control Boost Converter Under current mode control, iL1 is fed back when Q1 is turned on to determine the on-time of Q1 by comparing it to a current control signal iC. A compensation ramp of slope -mC is normally added to avoid sub-harmonic oscillation. Figure 2 shows the current waveform of an on period. The averaged state equation is as follows: Figure 2. Inductor Current Waveform at the On Period iL1 = iC - mCdTSW - m1 2 dTSW, (19) where m1 = QIN L1 (20) is the slope of iL1 during the on period. By adding small signal perturbations to the above equation, T ~ ~ ~ ~ ~ IL1 + iL1 = IC + iC - mC(D + d)TSW - SW (M1 + m1)(D + d). 2 (21) By applying the linearization technique (assume that the high order non-linear terms are small and negligible), a set of DC and AC equations can be obtained as follows: DC equation: IL1 = IC - mCDTSW - TSW M1 D 2 (22) where M1 = VIN L1 AC equation: ~ ~ ~ T ~ T ~ iL1 = iC - mCTSWd - SW M1d - SW Dm 1 2 2 (23) Define T2 = TSW , 2 (24) TSW (2mC + M1) TM = 2 (25) From (20), (23), (24), (25), ~ Q ~ ~ ~ iL1 = iC - TMd - DT2 IN . L1 (26) Substitute (13) into (15), ~ VIN . ~ ~ sL1iL1 = ~ QIN - (1 - D)Q OUT + d (1 - D) 4 AN-1994 Modeling and Design of Current Mode Control Boost Converters (27) SNVA408B – January 2010 – Revised April 2013 Submit Documentation Feedback Copyright © 2010–2013, Texas Instruments Incorporated Modeling of a Current Mode Control Boost Converter www.ti.com Substitute (27) into (26), ~ d= ~ ~OUT - 1 + sL1DT2 ~ QIN sL1iC + (1 - D)Q L1 . VIN + sL1TM (1 - D) (28) By substituting (28) into (18), the small signal model of the current mode control boost converter can be formulated as follows: ~ + G (s)i~ GNC(s)Q IN IC C ~ , QOUT = '(s) (29) where GNC(s) = ROUT(1 - D)(1 + sRCOUTCOUT) ^(1 -VD)T M IN + DT2 sDT2 1 + ROUT(1 - D)2 ROUT(1 - D)2 L1 ` GIC(s) = ROUT(1 - D)(1 + sRCOUTCOUT) 1 - s '(s) = 2 + ROUT(1 - D)2TM ^L +s 1 L1 ROUT(1 - D)2 (1 - D) VIN + RCOUTROUTCOUT(1 - D)2 TM + s2 L1COUT (ROUT + RCOUT)TM (1 - D) VIN + (ROUT + 2RCOUT)COUT ` (1 - D) VIN If the current iL1 is sensed by a resistor RSN connecting between Q1 and the ground, the current control signal iC can be converted to a voltage control signal νC. The relationship between the output voltage and the voltage control signal can be formulated as follows: GIC(s) ~ ~ QC , QOUT = '(s)RSN (30) SNVA408B – January 2010 – Revised April 2013 Submit Documentation Feedback AN-1994 Modeling and Design of Current Mode Control Boost Converters Copyright © 2010–2013, Texas Instruments Incorporated 5 Principle of a Lag Compensator 4 www.ti.com Principle of a Lag Compensator Figure 3. Frequency Response of a Lag Compensator A lag compensator consists of a pair of pole and zero at the frequency fPC and fZC, with fPC < fZC. It also provides a dc gain AC. As shown in Figure 3, the lag compensator provides an attenuation in magnitude at the high frequency. The degree of attenuation is determined by the distance between fPC and fZC. It is because the magnitude is decreased at a slope of 20dB/decade between fPC and fZC. The lag compensator also provides a phase lag. However, fPC and fZC can be placed at a low frequency (much lower than the frequency of interest, for example, the cross over frequency fC) such that the lag compensator nearly does not affect the phase at the high frequency. The aim of designing a lag compensator is to provide a desired phase margin for the compensated system. Starting from a bode plot of an un-compensated system, and a requirement of phase margin of Φm, a new fC can be selected at the frequency corresponding to 180° - Φm of the un-compensated system. Then the magnitude of the un-compensated system at fC is found. The magnitude at fC can be attenuated to 0dB by the lag compensator through proper design of fPC and fZC. As a result, the compensated system will have a phase margin of Φm, and the cross over frequency will be fC. An illustrative example (see Section 5) will be presented to show the design steps. Figure 4. A Lag Compensator Implemented by a Transconductance Amplifier Circuit A lag compensator can be implemented by a transconductance amplifier, with an open loop gain of gm and an output impedance of R0, connecting to a resistor RC1 and a capacitor CC1 in series to the ground, as shown in Figure 4. Let the negative input of the amplifier is connected to a reference voltage VREF, and the positive input is connected to the output voltage νOUT through a resistor divider network implemented by RF1 and RF2, the transfer function relating νC and νOUT is QC = RF2 1 QOUT - VREF gm R0 // RC1 + SCC1 RF1 + RF2 (31) By adding small signal perturbations, the AC equation can be obtained as follows: a QC = RF2 RF1 + RF2 gmR 0 1 + sRC1CC1 1 + s(RC1 + R0)CC1 a Q OUT. (32) Hence, 6 AN-1994 Modeling and Design of Current Mode Control Boost Converters SNVA408B – January 2010 – Revised April 2013 Submit Documentation Feedback Copyright © 2010–2013, Texas Instruments Incorporated Illustrative Example www.ti.com RF2 AC = 5 RF1 + RF2 gmR0, fPC = 1 , 2S(RC1 + R0)CC1 fZC = 1 . 2SRC1CC1 (33) Illustrative Example The design of a current mode control Boost converter with a nominal input voltage of 5V and an output voltage of 12V and an output current of 0.5A will be shown. The major components are listed in Table 1. A current mode controller LM3478 will be used. The parameters of the LM3478, which can be derived from the data sheet, are also listed in Table 2. Table 1. Major Parameters of the Example Boost Converter Parameter Value VIN 5V VOUT 12V ROUT 24Ω L1 10 µH COUT 150 µF RCOUT 0.05Ω fSW 400 kHz RSN 0.05Ω RSL 604Ω Table 2. Parameters of the LM3478 Parameter Value VREF 1.26V gm 800 µΩ-1 R0 AV/gm = 38/800 µΩ-1 = 47.5 kΩ VSL 92 mV Other parameters of (30) are calculated below. From (13), D = 0.5833 From (24), T2 = TSW 2 = 1 2fSW (34) (35) T2 = 1.25 µs The parameter mC is determined by an internal compensation ramp VSL and an external compensation ramp determined by an internal current of 40 µA passing through an external resistor RSL. It can be calculated by the following equation: mC = (VSL + 40 µA x RSL)fSW/RSN = 929280As-1 (36) From (25), TM = VIN TSW 2mC + L1 2 = 2.9482A (37) SNVA408B – January 2010 – Revised April 2013 Submit Documentation Feedback AN-1994 Modeling and Design of Current Mode Control Boost Converters Copyright © 2010–2013, Texas Instruments Incorporated 7 Illustrative Example www.ti.com Hence, all parameters of (30) are obtained. A bode plot of (30) with the above parameters is shown in Figure 5. The DC gain, zeros, and poles are DC gain: 36.39dB Zeros: 53 kHz, 66 kHz (right half plane zero) Poles: 133 Hz, 65 kHz (38) (39) (40) Figure 5. Frequency Response of the Un-Compensated System The design of the lag compensator can be achieved by following (32). Since VOUT and VREF are 12V and 1.26V respectively, we can design that RF1 = 84.5 kΩ RF2 = 10 kΩ (41) (42) From (32), AC = RF2 g mR 0 RF1 + RF2 = 4.02 = 12.09 dB (43) In this example, a compensated system with a phase margin of around 90° is desired. From Figure 5, fC can be selected as 3.5kHz (the frequency at which the phase is around 180° - 90° = 90°). The attenuation required is 7dB + AC = 19.09dB, which implies that the distance between fPC and fZC should be 0.96 decade. Select fZC to be 350 Hz, i.e. one decade lower than fC, then fPC should be 38.3 Hz. 1/RC1CC1 = 2π x 350 Hz (44) 1 = 2S x 38.3 Hz (RC1 + R0)CC1 1 - R1CC1 R0CC1 = 2S x 38.3 Hz CC1 = 78 nF RC1 = 5.85 k: 8 (45) AN-1994 Modeling and Design of Current Mode Control Boost Converters SNVA408B – January 2010 – Revised April 2013 Submit Documentation Feedback Copyright © 2010–2013, Texas Instruments Incorporated Conclusion www.ti.com Figure 6. Frequency Response of the Compensated System with 90° Phase Margin Finally, select RC1 = 5.9 kΩ and CC1 = 100 nF. The frequency response of the compensated system is shown in Figure 6. It can be found that the 0dB point is at around 4 kHz, and the phase margin is around 95°. 6 Conclusion This application note details the modeling of an open loop and a current mode control boost converter under the continuous conduction mode. The principle and design of a lag compensator have also been addressed. An example has been presented to illustrate the design. A lag compensator has been designed for a compensated system with around 90° phase margin. The selection of a desired phase margin affects the transient response of the output voltage. Moreover, some practical systems are suffered from noise, and transient responses are not a major concern. A lower cross over frequency may be required. In this case, the application of the dominant pole compensation method may be more appropriate. The lag compensator can be easily changed to a compensator with a dominant pole by setting RC1 to zero, that is, to eliminate the zero. Application engineers are suggested to design properly based on practical situations. 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